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3590 East Columbia St
Tucson, AZ 85714
520-628-7415
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A Compact Nested High Voltage Generator for Medium Pulse
Duration Applications
R. J. Adler, J. Gilbrech, K. Childers, E. Koschmann
Applied Energetics
Abstract
The “Nested High Voltage Generator” (NHVG) topology
is an effective way of producing and grading high DC
voltages. It has been applied to a variety of technical
problems including semiconductor ion implantation, X-ray
security, and electron beam irradiation. We have built a unit
for pulsed power applications including such applications as
pulsed X-ray generation, pulsed plastics’ processing,
medium power microwaves, and pulsed ion beam annealing.
This unit is designed to produce 250 kV and up to
5 amperes for pulses of up to several milliseconds. Previous
pulsed versions of the NHVG used “hard tube” power
systems, but this unit uses series resonant solid state drive.
Repetition rates will vary for this machine from 1 pps to
1 kHz depending on the applied pulse format. We will
report on performance and prospects for higher power
operation.
forming network can also be used leading to the requirement
for higher insulating voltages than operating voltages.
In many applications the pulses are long enough so that
the amount of energy storage required at high voltage is
unacceptable. Alternately capacitive energy storage is
presently much smaller at low voltage than at high voltage.
In those applications, the capability of the accelerator as a
direct pulsed power supply becomes important. For
example if a beam of 10 A at 500 kV is required for a
millisecond, it requires 5 MW and 5 kJ. The 5 kJ can be
supplied by a modest “supercapacitor” capacitor bank but
will be bulky and expensive if created from a set of 100 kV
capacitors.
We have studied the use of our “Nested High Voltage
Generator” technology1 for this class of application. In
these applications the intrinsic capability of the power
supply is the critical question.
II. THEORY
I. INTRODUCTION
At energies of 100s of kV and intermediate currents
(amperes), pulse compression is often achieved by using a
grid controlled ion or electron beam to discharge the
capacitance of an accelerator to make a pulsed beam1. This
has been used in applications such as Free Electron Lasers,
accelerator injectors, grid controlled microwave tubes and
other applications with considerable success.
DC and quasi-DC HV power supplies use transformers,
voltage multipliers, diode stacks, and other components to
produce power at a high voltage. Voltage multipliers have a
maximum power output. A typical voltage multiplier
running at 50 kHz and 50 kV RF input with 400 pf
capacitance has the power output as shown in Figure 2.
Multiplier Outputs
500
450
400
Voltage (kV)
V(4 Stage)
350
P*10(4 Stage)
300
V(3 Stage)
P*10(3 Stage)
250
V(2 Stage)
200
P*10(2 Stage)
150
V(1 Stage)
P*10(1 Stage)
100
50
0
0
200
400
600
800
1000
Current (mA)
Figure 2. Voltage Multiplier Outputs.
Figure 1. NHVG Operational Diagram
These techniques are often limited by the energy storage
capabilities of the accelerator or other system which is used
to provide the voltage. If a pure high voltage capacitance is
used as the energy storage medium, there can be a
significant droop in the pulse when loaded. A pulse
The power output of (say) a 4 stage multiplier is limited
to 20 kW for our parameters. Single stage multipliers allow
us to reach higher powers but they are clearly not practical
above 200 kV due to the large primary voltages required.
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3590 East Columbia St
Tucson, AZ 85714
520-628-7415
http://www.appliedenergetics.com/highvoltage.asp
Charging the single multiplier is the challenge and the
NHVG architecture is well suited to that challenge.
A magnetic core can be used to provide power for HV
systems, but conductive cores are awkward to insulate (for
example the Insulated Core Transformer or ICT) or they
must be non-conductive as in a non-conductive ferrite.
A “dynamitron”2 configuration can be considered for high
powers but the structures tend to become large for such
powers independent of the average power. The reason is
because they are capacitively coupled, the total voltage is
applied across the capacitor.
We have investigated the use of the Nested Generator as a
direct drive power supply at high voltage and >1 MW
powers3. The nested generator consists of concentric nested
conductors separated by insulators. Each pair of conductors
has a power supply internal to them. So for N+1
conductors, there are N power supplies and these power
supplies are in series. In general we have built these units as
“air core” units with no magnetic material. We power the
unit with parallel or series resonant circuit which creates
axial magnetic flux through a solenoidal primary coil. The
power supplies are powered by coils which have a voltage
proportional to the rate of change of magnetic flux times the
area-turns product.
We wished to investigate the general properties of such
geometries for power transfer. In general we operate the
units with resonant circuits where we can readily remove
2/3 of the energy in the magnetic field. The total energy
“recirculated” in the magnetic field is the primary inductive
energy 0.5LI2 times the frequency times 2 (for each
direction of field) = fLI2. For example if we wish to drive
500 kV and 5 Amperes (2.5 MW) at 100 kHz we require a
primary inductive energy of at least 2.5 MW/2/100 kHz =
12.5 Joules. This can be produced (for example) with a
4 uH coil at 2.5 kA with 100 % of the energy extracted. In
practice the energy extracted is limited to the energy in the
volume of the secondary and so is approximately kfLI2
where k is the coupling coefficient. Note that this is not an
absolute limit but rather it is a practical design rule.
The multiplier relationships in Figure 2 tell us that the use
of voltage multipliers in these geometries will limit the
power, and so we have used two series half wave rectifiers
per stage in order to maximize the available power.
Either series or parallel resonance can be used for the
primary circuit, but it is quite simple to produce high
voltages and currents simultaneously in series resonant
circuits. For that reason the experiments described here are
those on series resonant circuits.
III. SYSTEM DESIGN
A. Design Parameters
Handling over a megawatt of instantaneous power is a
significant design task. Table 1 illustrates expected currents
in each subsection of the NHVG. As one can see the current
reaches large values on the left hand side to allow for a large
setup in voltage. As such it is important to not only pay
attention to fusing currents but also basic AC impedances.
A wire might have a DC impedance of a few milliohms,
however due to the skin effect, an instantaneous current
pulse may have an impedance orders of magnitude higher.
That, in turn, can lead to extremely large amounts of
instantaneous power which have to be dissipated.
Location
Primary
Resonant
Simulated
Currents
Voltage
Est. Power
Loss*
6000A
8000V
3600W
Secondary
15A
12500V
20.25W
Output
Rectifiers
15A
25000V
54W
*Power Loss in parasitics present in subsection over 1mS pulse at
repetition rate of 10 Hz
Table 1. Estimated Power Loss per section
The system therefore has to handle the high current and
loss on the primary side. The secondary side ends up being
quite a bit less lossy because the secondary RMS current is
relatively low. In order to optimize the efficiency while
being conscious of the skin depth constraints, we built the
primary with a copper foil. The winding will be composed
of foil that is half of the skin depth at the operating
frequency. The width of the foil still results in a large crosssectional area for the primary coil. Our design goal for the
primary was to have the overall AC resistance of the coil at
operational frequency to be 5 milliohms or less (30 V
resistive drop).
Figure 3. System Assembly 3D
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3590 East Columbia St
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520-628-7415
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B. Inverter Design
F. Multiplier Design
The inverters used in the system were quad H-bridge
inverters utilized on numerous previous projects by AE.
These inverters were designed for 50 kHz maximum
frequency but for test purposes we elected to operate them
as high as 130 kHz. The IGBT losses were large, but given
the low duty cycle and active cooling the system performed
adequately. These systems have been heavily ruggedized
and are capable of driving into full arc conditions with no
damage suffered. For future projects that involve high
power transfer requirements for pulsed applications a
MOSFET based drive would be implemented. This type of
drive would be better suited for the high resonant frequency
and current sharing aspects of the system.
The multiplier pucks house the secondary windings,
storage capacitance, diode rectifiers, and/or bipolar series
multiplier diodes. Each puck contains 9.4 nF of storage
capacitance. This allows for 48.95 Joules of energy stored
at the peak output voltage. This energy storage allows for
the system to respond instantly to power draw while the
primary drive resonance cycles up to full voltage. A full
wave rectifier scheme was utilized to convert the resonant
AC drive to a DC output voltage. The rectifier board was
designed such that it could be changed easily to a bipolar
series multiplier for future systems.
Multiplier spacing is at 30 kV/in. The multiplier board
has twelve devices in series to allow for full voltage holdoff, ripple voltage when utilized as a series voltage
multiplier, and also instantaneous voltages caused by
subsection arc events. The devices are spaced such that the
components have .5 inches distance from their nearest
neighbor which is 6 kV different in potential. This gives us
a significant design safety factor on the multipliers.
C. Foil Carrier/Strongback Design
The strongback is the part of the system that has the
Kapton and copper foil wrapped upon it. The multiplier
assembly and accelerating column nests inside of this
structure. It is responsible for grading the axial electric field
and also establishing an even magnetic field throughout the
internal NHVG structure. The insulating foil used 100 mils
of 5mil Kapton. Kapton has a dielectric strength of 3,900
volts/mil as per ASTM-D149-64. We’re utilizing 100 mils
of Kapton to insulate 50kV, thus our volts/mil is 500V/mil.
Historically previous successful operating systems have
used this same amount of solid material for insulation.
D. Primary Design
Figure 4. Multiplier Puck Assembly
The Primary voltage was designed to 8-10kV. Primary
windings were spaced via 5 mil Kapton film. For the 6 turn
primary that means we will have a volts per turn of
1666.66V. The insulation of the of the Kapton foil wire will
hold off 3,900V. The design margin in the 6T primary is
2.34X more than needed.
Initial estimations and
simulations denoted approximately 6kA on the primary
during the output pulse. The final primary AC resistance
measured during testing was 10 milliohms.
E. Secondary Design
The secondary windings were composed of four layered
windings. These windings were three layers of 12 turns of
20 AWG magnet wire wound with an insulating layer of
Kapton between the layers. Since the secondary voltage is
12.5 kV per winding the volts/turn on the total 36 turns was
347 V. Since we have two layers sitting on top of each
other the second layer will at the worst point see the 4.16 kV
differential voltage. 30mil of Kapton was utilized between
layers along with careful winding techniques to ensure no
breakdown occurred in this area.
G. Output Section Design
The output section was designed to accept two forms of
power delivery. The primary design was for an integrated,
removable electron gun and associated accelerating region
that is common to most NHVG units. The second option
that was designed was to connect to a 250kV X-ray
connector. This secondary option would allow the NHVG
to operate solely as a voltage source and or allow the
electron gun to be located away from the voltage/filament
source. These options are collocated in this single design,
the only modification necessary to switch between the
options are an adapter flange for the output end.
H. Accelerating Column Design
The accelerating column and cathode design are an
integral assembly. This assembly is designed to operate in
vacuum and is sealed such that it resides nested within the
oil volume of the NHVG. The chosen cathode is an off the
shelf part from Kimbal Physics, ES-440. The accelerating
column is composed of a Rexolite tube machined to hold a
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3590 East Columbia St
Tucson, AZ 85714
520-628-7415
http://www.appliedenergetics.com/highvoltage.asp
number of grading rings, as shown in figure 3. These
grading rings step the voltage down in increments of 50 kV.
This allows for a gradual voltage grading that puts the
vacuum connection at ground potential and also an
accelerating region for the electron beam.
Figure 5. Accelerating Column Assembly.
I.
Final Build
Final system assembly went well. Some modifications to
the strongback design were needed to ease manufacturing
concerns. The most difficult and time consuming aspect of
the assembly process was cutting then winding the
Kapton/Copper foil layers onto the strongback piece. In the
future this process can be greatly simplified by ordering
Kapton and copper foils cut to width and length. Figure 6
illustrates the system as built, after the final test run. In this
image the multiplier stack has been pulled out for ease of
viewing.
allowed for changes to be checked before investing time and
effort into the modifications.
As shown in figure 7 the NHVG was capable of a 250kV
output voltage in to an 83.3 kOhm load resistor. The
channel two waveform shows the voltage on the last resistor
in a resistor bank composed of 35 equal resistors in series.
This represents an instantaneous power of 0.75 MW.
Output at 250kV ended up being limited to 3A due to the
IGBT limitations. Our budget only allowed for four inverter
boxes to be constructed. Each inverter box was limited to
1600 A of resonant current. With the addition of further
inverters the system would be expected to operate above
1.5 MW of instantaneous power without difficulty. The
waveform shown was generated by pulsing the system up
from a zero voltage state. In true operation, the response
time would be limited by the grid circuitry associated with
the electron gun. One can see that the system responds to
full voltage in approximately 200µS into fully loaded
circumstances.
Future work will involve integrating the accelerator
column with the rest of the accelerator and DC operation at
up to 15 kW average.
Figure 6. Final System Build
IV. TESTING
System
performance
demonstrated
remarkable
efficiencies at high loading, 40k Ohms and 50k Ohms
resulted in efficiencies over 80%, while operation in the
80k-150kohm regime performed over 70%. It should be
noted that no effort was expended on optimizing the main
source of loss (the use of IGBTs rather than MOSFETs). In
future designs the inverters will have MOSFET inverters
designed for operation above 100 kHz.
Simulations performed allowed for an extremely high
confidence in modifying the system. As shown in figure 7
the system responded almost identically in simulation and in
testing. This attention to detail in our simulation modeling
Figure 7. Output Waveform 250kV at 3 Amps (Simulated Versus
Experimental)
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3590 East Columbia St
Tucson, AZ 85714
520-628-7415
http://www.appliedenergetics.com/highvoltage.asp
VI. REFERENCES
V. CONCLUSIONS
We have designed and constructed a dual operation
capability Nested High Voltage Generator in a rapid
prototype research and development program. This NHVG
is designed around a modular approach that allows for
future designs in the 100kV to 600kV voltage range and 0.5
to 5 MW peak power regimes. These supplies are capable
of integrating in a nested electron gun or simply functioning
as a pulsed or DC high voltage power supply.
[1] R. J. Adler and R. J. Richter-Sand in proceedings of the
IEEE Pulsed Power Conference 1991, p. 92. IEEE
CH3180-7/92.
[2] M. R. Cleland “Voltage Multiplication Apparatus” US
Patent 2,875,394.
[3] R. J. Adler, Patent Pending.
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